Sp138-35 Energy Absorption FRP Reinforced-beams
Transcript of Sp138-35 Energy Absorption FRP Reinforced-beams
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Synopsis,
SP 138-35
Flexural Behavior and Energy
Absorption o Carbon FRP
Reinforced Concrete Beams
by T. Kakizawa S. Ohno
and T. Yonezawa
Research and development ofFRP bars and cables for reinforcements of
concrete structure has recently been carried out. The basic behavior of the concrete
members reinforced with these FRP bars has became well understood. However,
there are still
debatable
points in terms of the
design concept
such as the
recommended failure mode or required toughness and ductility. The authors
carried out loading tests of the 6 concrete beams reinforced with carbon FRP bars
and cables in order to discuss the both serviceability and ultimate limit states. The
specimens includes
the RC, PC, PPC
members.
The main factors are bond
properties of the FRP reinforcements and prestress force. The experimental results
show that cracking and deformation behavior vary with the prestress force and
bond property of FRP bars, and that the reasonable serviceability condition will be
achieved by controlling these factors. Also, the failure mode were affected by
these factors and the reinforcing systems, despite these specimens have almost
same reinforcement ratio. In relation
to
the failure mode, the energy absorption,
which is defined as the area enclosed by load-deflection curve, was measured to
discuss the toughness and ductility for the ultimate limit state. The authors
recommend that the design should take into account the toughness based on the
energy absorbed before the maximum load.
Keywords: Absorption; beams supports); cable; carbon; cracking
fracturing); deformation; ductility; failure; fiber reinforced plastics; flexural
strength;
prestressed
concrete; reinforced
concrete
585
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586 Kakizawa Ohno nd Yonezawa
Tadahiro Kakizawa, is a research engineer in Takenaka Research Laboratory. He
received an MS in civil engineering from the University
of
Tokyo. He is currently
working in the area
of
development
of
new structural materials.
Sadatoshi Ohno, is a senior research engineer in the advanced materials group
in
Takenaka Research Laboratory. He received his Ph. D. from the University
of
Sur
rey, U.K. His research interests include fracture mechanism, alkali aggregate reac
tion, fiber reinforced composites, and new structural materials.
Toshio Yonezawa,
is
a chief research engineer in the concrete materials group
in
Takenaka Research Laboratory. He received his Ph.D. from the University of
Manchester Institute University, U.K He has been extensively involved with re
search on corrosion problems
of
steel
in
concrete, high strength concrete, fiber
reinforced concrete and new materials in construction field.
INTORODUCTION
Substantial effort have recently been made to develop fiber reinforced
plastics FRP) bars and cables for reinforcement
of
concrete structures. There
is
great interest
in
the high-strength, rust-free, and non-magnetic properties
of
such
new materials.
With
regard to the design
of
structural members using RP
reinforcement, it has been reported that flexural behavior can be predicted based
on conventional flexural theory for reinforced concrete. However, the members
reinforced with
RP
bars or cables exhibit brittle failure prope11ies since FRP
materials have no plastic region, while conventional reinforced concrete and
prestressed concrete show a ductile failure behavior because of the yield of the
steel reinforcement. From this viewpoint, an appropriate design method for
ultimate limit states
of
concrete members reinforced with FRP still remains
to
be
investigated.
In
related discussion, it has also been reported that the compression
failure mode is preferable for such RP reinforced concrete members, because the
failure
of
the member proceeds more gradually
at
the ultimate state compared with
failures
of
those governed by brittle FRP breakage I).
In
contrast, another opinion
is that alternative design methods which can allow for brittle failureof members
due to FRP breakage should be considered for reasonsof economy and rationality
2).
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FRP Reinforcement 587
On the other hand, various studies have worked to improve the ductility
of
FRP reinforced concrete by controlling bond properties
of
the FRP
reinforcement
or
placing the
FRP
reinforcement in multiple stages 3). Also,
attempts on improving brittle behavior by constra ining the compression zone
of
the reinforced members have been reported 4), 5).
However, the important concern is to secure the required ductility both for the
members and the structures being designed, and in order to do this more thorough
discussion
of
the appropriate design needs
to
be undertaken.
EXPERIMENTS
In this experiment, small beam specimens
of
rectangular section were
adopted as shown in Figure I and reinforced concrete RC), prestressed concrete
PC), and partially prestressed concrete PPC) systems using FRP reinforcement
were tested. Cable strand of carbon fiber reinforced plastics CFRP) were used as
prestressing tendons, and two kind
of
tensile
reinforcement- CFRP
cable strands
and CFRP deformed bars- were used. Tables I and 2 give the physical propetties
of the reinforcing materials and the strength
of
the concrete used, respectively.
Loading tests
were
carried
out on
16
types
of
specimens
with different test
parameters - prestress force, reinforcement type, bonded
or
unbonded tensile
reinforcement, and prestressing cable
as
shown in Table 3. The sectional areas
of
FRP reinforcement given in this table are the nominal cross sectional area
including the resin. Specimen No. I is an ordinary reinforced concrete beam
incorporating deformed steel bars, specimen No. 2
is
an RC beam using FRP
reinforcement
specimens No. 3
through
6
are PC
beams
without tensile
reinforcement, and all
other
specimens are
PPC beams. Specimen
No.
16
although made of the same material as specimen No. 13, was made with a 5 mm
thick permanent form reinforced with polypropylene fiber net to improve in
service propet1ies. Unidirectional loading was applied to all beams, which have a
span
of
170
em
and a moment span
of
30 em. n the tests, load, deflection, strain in
the concrete and reinforcement, and crack width were measured.
RESULTS OF EXPERIMENT ND DISCUSSION
Cracking and Deformation Properties
Table 4 shows the
results of the
loading
tests.
Reasonably
close
agreement was obtained between the measured and calculated values of cracking
load. Figure 2 illustrates the cracking patterns of the loaded beams. Provided that
the service load is about
one
third
of
the maximum load, no appreciable cracking
was recognized in the
PC
and
PPC
specimens and the cracking was very fine even
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588 Kakizawa, Ohno, and Y onezawa
when it did occur. The cracks in specimen No.2 are very small, less than 0 1 mm,
at the service load and it is thought that no serious problems would arise in an
actual application as far as cracking is concemed. However, since the specimens
used here were small, it must be taken into consideration that cracks tend to be
smaller than in actual concrete members.
The distribution
of
the cracks along the beams differed according to the
specimen. When the specimen has no tensile reinforcement in the PC member
specimens No. 3 through 6) or has a partially unbonded tensile reinforcement in
the PPC members, fewer cracks were observed. In the case
of
the unbonded PC
specimen CPC58U), cracks were particularly concentrated in the moment span.
When the working load becomes high over
13
kN) in this specimen, the
deformation is concentrated only at the center, as demonstrated by the deflection
distributions shown in Figure 3. This may cause local secondary stress at the
deformed area and/or frictional damage contacting with the sheath. These effects
are not desirable because FRP reinforcement may break earlier than expected.
On the other hand, specimens with CFRP deformed bars used as tensile
reinforcement show good crack distributions, and have closer crack spacing than
conventional RC members. However, longitudinal splitting cracks were found
along the reinforcement at the ultimate state. These cracks were related to the
dimensions of the specimen, the concrete cover, and the bond properties of the
reinforcement. The bond properties of FRP reinforcement are greatly affected by
their configuration
of
deformation, and this remains an area for further study.
In
specimen No.
16
CPRC38UB-NET), where the permanent form
reinforced with
polypropylene fiber
net was
used, the
cracks were
finely
distributed at a spacing ranging from a few millimeters up to one centimeter,
although these cracks are not illustrated in this paper. This behavior is
advantageous when cracking in the application must be limited, and when the
design calls for a wider range of service conditions.
Ultimate Load and Failure Mode
Figures 4 a)- f) show load-deflection curves for the specimens. The
results for specimens reinforced with FRP differed depending on the type of
reinforcement and the differences in bonding. The obtained curves are not
basically different from those
of earlier reports. When the results for CPRC24BB
YY are compared with those for CPRC24-
YR,
CPRC38BB-YY with
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RP Reinforcement 589
CPRC38BB-YR, and
CPRC38UB-
YY with
CPRC38UB
the ultimate load is
found to be
15
to 20 higher for specimens using CFPR deformed bars rather than
CFRP
cables
as
the
tensile
reinforcement in spite of
the
almost identical
reinforcement system and same reinforcement ratio. The reason for this difference
is thought to be due to be the bonding characteristics of the reinforcement. When
two kinds
of
reinforcement with different bond properties are used simultaneously
in the specimen, the actual working stress may be different from the prediction,
which is based on the assumption that plane sections before bending remain plane
after bending.
The calculated and experimental
values
of ultimate strength
were
compared in
Table
4.
The
calculated ultimate strength was derived from the
requirement
of
strain compatibility and equilibrium
of force
by repeating
calculation for the divided elements
of
the beam section. In this calculation, the
relationship between concrete stress and strain was assumed to be expressed by
Umemura's equation(6), as follows.
0
=
O cu
{ 6.75 ( e (-0.819 e ( -1.218
where =_ _
Ecu
cr
concrete stress,
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590 Kakizawa Ohno
nd
Y onezawa
and the arrangement of prestressing cables and reinforcement.
The failure modes predicted by calculation and the results observed from
the experiments are given in Table 4. Although they agree relatively well, there is
a difference between predicted and experimental results for PPC members with
unbonded prestressing cables. Although the reason for this is not clear, some local
stress may have been induced because the measured strain in the prestressing
cables was less than the nominal failure strain at the time of fracture.
According to earlier work, the compression failure mode is slightly
ductile compared with the reinforcement failure mode in FRP reinforced concrete.
However, in this experiment, no great difference could be seen even in the case of
a compression failure. This is because the FRP reinforcement failed during
compression failure when the reinforcement ratio was close to the balanced failure
state CPC69B and CPC58B) See Figure 4). Considering these points, additional
reinforcement over the amount required to obtain compression failure needs be
incorporated in
order
to ensure a compression failure without
FRP
failure.
However, this still presents problems in terms
of
economical design. t is also
difficult to specify the failure mode in the design, since this would mean taking
account of changes in the material properties over the whole lifetime and
of
the
scatter in fracture strength of the FRP reinforcement.
n
the case
of
PPC members
with
FRP
cables as tensile reinforcement, on the other hand, the beam specimens
deformed by relatively large amounts even after failure of the prestressing cable.
This shows the possibility
of
designing FRP reinforced concrete members with
such deformation behavior by controlling the amount of reinforcement and the
bonding properties.
Energy Absorption
n
terms of design, the ductility required of a structural member should
vary depending on its type, importance, service conditions and so on.
n
the design
for conventional reinforced concrete, the brittle failure of members has been
avoided considering safety. Therefore, normally designed reinforced concrete for
flexural members are ductile, because their energy absorption is due to the capacity
of the steel to deform; that is, they have adequate ductility and great energy
absorption.
n the case of FRP reinforced concrete members, avoidance of the brittle failure
may not be easy and economical. Also, the ductility factor which is usually
expressed as the ratio of the ultimate deformation to the deformation at first yield is
not considered to be proper to assess the characteristics of FRP reinforced
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RP Reinforcement
59
concrete. The ductility factor is a index to express the deformation capacity and
consequently shows the energy absorption. Therefore evaluation of energy
absorption would be very important in the design of FRP reinforced concrete,
although a discussion
of
the proper safety factors has to be continued.
Table 4 and Figure 5 show the absorbed energy, which is defined to be
the area enclosed by the load-deflection curve for each specimen. The energy
absorbed before and after the maximum load is shown separately. The values of
the total energy absorption are unlikely to be affected by the failure mode within
the range of this experiment s conditions. PPC members tended to indicate
greater energy
absorption
than PC despite having the same amount of
reinforcement. This may imply an advantage for PPC. When the absorbed energy
after the maximum load is compared, the PC members show no energy absorption
after failure
of
the
FRP
cable at the ultimate load because only prestressing cables
were placed in the PC members in this experiment.
On the contrary, the unbonded PC specimen CPC58U, which failed in
compressive mode, showed the same energy absorption before the maximum load
as after the maximum load. In PPC members, some energy is absorbed even after
the prestressing cables have failed, since FRP reinforcement could still sustains a
load; it thus allows for further deformation. Also in the case
of
PPC members
using FRP reinforcement and prestressing cable of different bond prope11ies, the
amount of absorbed energy after the maximum load tended to be higher when
CFRP cables were used
as
tensile reinforcement, while the energy absorbed before
the maximum load was higher when CFRP deformed rods were adopted
as
tensile
reinforcement. Thus it is possible to obtain various energy-absorption prope11ies
by controlling the reinforcing system. However, evaluating the energy absorption
after the maximum load is technically difficult (The theoretical calculation is
thought to be possible, but there are some problems in accuracy. ) If the concrete
members are such that energy absorption is not expected, i.e. only vertical loads
act and the member doesn t need resist the earthquake load, it may be meaningless
to evaluate the energy absorption over such a range in the design.
The energy absorption
of
FRP reinforced concrete beams and slabs
under the influence of vertical forces should be evaluated by the total energy
absorption up to the maximum load. In the case of the members where an
evaluation of repeated energy loads, such as earthquake loads, is required, fUI her
detailed studies will be necessary.
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592 Kakizawa Ohno
nd
Y onezawa
CONCLUSIONS
In this study, the cracking behavior and failure properties and the energy
absorption of FRP reinforced concrete have been investigated experimentally,
with the prestress force and bonding properties of the FRP reinforcement taken as
the experimental factors. The failure mode and deformation behavior are found to
change according to the reinforcing system. The absorbed energy s affected by the
reinforcing system, but little by the failure mode, within the range of these
experiments. PPC members absorb more energy than PC in spite
of
the same
amount of reinforcement. Based on these results, design criteria were discussed n
connection with energy absorption and failure mode. t is recommended that the
design should take into account the ductility evaluated for the energy absorbed
before maximum load.
REFERENCES
I) H.Mutsuyoshi, A.Machida, and K.Uehara, Mechanical properties and
design method
of
concrete members reinforced by Carbon Fiber Reinforced
Plastics, Proceedings of the Japan Concrete Institute, 12-1, pp. 1117-1122,
1990.
(2) H.Nakai, K.Mukae, H.Asai, and S.Kumagaya, Analytical study on bending
ultimate state of prestressed concrete beams with FRP rods, Proceedings of the
Japan Concrete Institute, 13-2, pp. 749-754, 1991.
(3) Y.Yamamoto, H.Maruyama, K.Shimizu, and H.Nakamura, Fractural
properties of concrete members with a multi-stage arrangement of CFRP, Japan
Society
of
Ci vii Engineering, Proceedings of the 46th Annual Conference, pp.
238-239, 1991.
(4) M.Odera, T.Maruyama, and Y.Ito, Improvement n compression failure
mode of
RC beams using CFRP rods, Japan Society
of
Civil Engineering,
Proceedings of the 46th Annual Conference, pp. 242-243, 1991.
(5) H.Taniguchi, H.Mutsuyoshi, A.Machida, and T.Kita, A proposal of
Improvement n failure mode
of
PC flexural members using FRP, Japan Society
of Civil Engineering, Proceedings of the 46th Annual Conference, pp. 244-245,
1991.
(6) Umemura, Uitimate strength and plastic behavior of reinforced concrete,
Transactions of AIJ, 1951.
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No
1
2
3
4
5
6
7
8
9
10
11
12
13
14
15
16
FRP Reinforcement
593
TABLE MECHANICAL PROPERTIES OF CFRP REINFORCEMENT
Nominal Ultimate
Elastic modulus
Type
Strength
(kN)
(GPa)
Carbon
FRP
96 (
10.5}
140
Strand cable
57 ( t 7.5)
Carbon
FRP
31 (
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594
Kakizawa, Ohno, and Yonezawa
Ctacking
Name of
load (kN)
No
~
pecinens
Calc.
I &SO 5.1
4.2
2CA::
4.1
4.2
3
CPC69II
12.4
13.4
4 IXS8B
12.3
11.9
s
a>c3llll
9.5
9.2
6 CPQi8U 10.4 11.9
~ Y Y
7.4
7.4
s ~ m
7.5 7.4
~ m
7.1
7.4
I O ~ y y
9.5
9.2
u p a m m
9.5
9.2
12 Cl fCB.B.YY
8.4
9.2
13 Cl fCB.B.m
8.0
9.2
14 CPfCllllli.YY
8.5
9.2
S
CPfCllllll.m
9.1
9.2
16,..,...,.........,
11.5
9.2
TABLE 4 TEST RESULTS
MaxinJm
Defteldion
nelgy
absorption
lctkm)
load (kN)
allhe
llliiiiSII8d
miXilun
oad
before altar
Calc.
II1IICirun
I Xi Tur
taal
value
mm)
load load
14.6 12.3 49.91 65.7>
65.7>
35.3 26.0
-
79.3 0.0 79.3
28.9
.25.7
21.99
50.3
6.9
5 7 ~
29.5 25.8 29.36 64.4 0.0 64.4
20.3 15.7 23.76 36.4 0.0
36.4
15.3 18.0 21.36 29.0 30.2 59.2
31.0
26.5
35.56
71.7 29.5
101.2
36.1 27.1 40.27 89.9 3.9 93.9
31.6
25.5
38.01 74.9 12.1 87.1
31.4 24.5 32.70 70.6 39.8
110.4
36.5
25.5
36.24 87.3
0.0
87.3
24.3
25.5
26.29 44.6
109.5
154.1
31.4
25.5
38.41 80.0 10.9
90.9
25.8 22.5 25.32 45.0 48.8 93.8
30.8 24.5 25.33 84.5 0.0
84.5
33.5 25.5 36.23 90 .4 4.5 94.9
I I 1 I I
I -
t 50 +
700
1000
Failure mode
Experimental
Calcurated
observation prediction
Yeild ol steel bals
Yeild of steel bals
Failn
d
IBnSie
ban;
Fabe
d
Tensile
IJus
B8iiiiiced
iiiiiure
Failure d PS
cabl8-
PS cable failure
Balanced
laiure
a11ar lalure
Failure
d
PS cable
Failure d
PS cable
~ l a i u r e ~ l a i u r e
~ l i u r e
~ f l i b
Failure ollensile bals
CorTpession
falJre
& CQIIllf8SSion
lalure
Failure ol PS cable
~ l a i u r e
ancllonsie bals
Failure ol
PS cable
FaiUe
of
PS
cable
and lansile bals
Failure
ol PS
cable
Balanced laiure
ancllansile bals
Falun of PS cable
~ l a i u r e
Balanced laiure
~ l a i u r e
Faiure of PS cable Failure
d
PS cable
Failure
of
PS cable FaiUa
of
PS cable
Faiure of PS cable
~ l a i u r e
100 .j
PC strand
CFRP
cable)
Fig. 1 Details of test specimens
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FRP Reinforcement
9
No.1 RC-SD
No.9 CPRC24UB-YR
I
Yl d{lliafj \ \
zs zs
I mrCwJh\ Y I
s zs
No.2 CRC
No.10 CPRC38BB-YY
I )
r
l\1 \\ r I
zs zs
No.11 CPRC38BB-YR
I r ~ \ I
zs zs
No.12 CPRC38UB-YY
r r)
t
zs zs
No.6 CPC58U
I
r
rhj 1
\\1 \J/
I
zs zs
No.13 CPRC38UB-YR
I c J d i ~ \ \ I
zs zs
zs zs
No.14 CPRC38BU-YY
No.7 CPRC24BB-YY
1cc
rflliYr \
zs
l
No.8 CPRC24BB-YR
Fig 2 Crack patterns of loaded beams
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596 Kakizawa, Ohno, and Yonezawa
0
-
5
E
10
c
1 5
J)
E
J)
20
)
~
Q_
25
0
30
- ~ - - - - - - - - . .
CFRC
+ + =
~ ~ ~ ~
3 5 ...........................T ' ' '(' '
-
*- CPRC38BB-YY
40 L _ ~ ~ ~ J _ ~ ~ ~ L ~ ~ ~ ~ ~ ~ ~ ~
0
42.5 85 127.5 170
Location em)
Fig. 3-Distribution of displacement
at
the load of
5
kN
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40r----------------------
z
~ 3 0
20
CRC
~
-
RC-50
10 20
3 4 5
60
eflection
mm)
a )
40r----------------------
~ 3 0
20
CPRC24BB YR
.../\
/
//_.
/.
r
~ / ~
CPRC24UB YR
CPRC24BB YY
O k ~ ~ ~ ~ ~ ~ _ J
z
~ 3 0
20
0 10 20
3 4
5 60
eflection
mm)
c )
CPRC38UB YY
C P R C 3 8 B U - Y Y ~ ~
O L ~ ~ ~ ~ ~ ~ ~ ~ ~ ~
0 10 2 3 40 5 60 7 8 90
eflection
mm)
e )
RP Reinforcement
597
40r----------------------
~ 3 0
-o
c
2
3 10
CPC69B CPC58B
CPC38B
/ /
... : ~
I
..
_ ; ; - - - - - - ~ - - - . . - -
CPC58U
O L ~ ~ ~ ~ ~ ~ ~
z
~ 3
0 10
2 3
40
5
60
eflection mm)
b )
O L ~ ~ ~ ~ ~ ~ ~
0 10 20
3
40
5
60
eflection
mm)
d )
40 r - - - - - - - - - - - - - - - - - - - - - - ,
z
~ 3
20
CPRC38UB YR
o ~ ~ ~ ~ ~ ~ ~ ~ ~
0 10 20 3 40 5 60
eflection mm)
f )
Fig. 4--Load-deflection curves
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98 Kakizawa Ohno and Yonezawa
0 20 40
60
80 100 120 140 160
Energy Absorption kN-cm)
Fig.
5 Comparison
of energy absorption